Driving apparatus for electric motor

ABSTRACT

The present invention relates to a driving apparatus which performs vector control based on an output current of an inverter. The driving apparatus of the present invention includes a vector controller ( 11 ) for transforming three-phase output currents of an inverter ( 10 ) into a torque current and a magnetization current, and controlling the torque current and the magnetization current. The vector controller ( 11 ) includes a torque-voltage control section ( 21 ) for determining a torque-voltage command value based on a deviation between a torque-current command value and the torque current, a magnetization-voltage output section ( 23 ) for outputting 0 as a magnetization-voltage command value, a target-magnetization-current determination section ( 26 ) for determining a magnetization-current command value based on a deviation between a torque-voltage command value and a target-output-voltage value, and a target-output-voltage determination section ( 27 ) for determining the target-output-voltage value.

TECHNICAL FIELD

The present invention relates to a driving apparatus for driving an electric motor, such as a synchronous motor or an induction motor, and more particularly to a driving apparatus which performs a vector control based on an output current of an inverter.

BACKGROUND ART

Commonly-used conventional methods for controlling a motor include a V/F control which involves outputting a voltage corresponding to a command frequency, thereby keeping a motor magnetic flux constant, and a vector control which involves decomposing an inverter output current into an excitation current and a torque current, and controlling the excitation voltage and the torque voltage so as to generate a motor current which is commensurate with a load.

The V/F control does not require a high-speed computation and can control a motor with a simple construction. However, the V/F control is poor in feedback information, and therefore high-efficiency control adapted for characteristics of each individual motor cannot be expected. Furthermore, since the V/F control does not detect a position of a motor rotor, a rotor of a synchronous motor can lose synchronism.

A sensorless vector control is a control technique which can prevent a synchronous motor from losing synchronism and can control the synchronous motor without using an expensive position sensor (see patent document 1). FIG. 19 shows a control block diagram illustrating the sensorless vector control. Three-phase currents Iu, Iv, Iw, detected by a current detector 12, are sent to a three-to-two phase transformation section 17, where the three-phase currents Iu, Iv, Iw on a stationary coordinate system are transformed into two-phase currents on the stationary coordinate system. The two-phase currents on the stationary coordinate system are sent to a stationary-to-rotational coordinate transformation section 18, where the two-phase currents are transformed, based on a phase θ, into two-phase currents on a rotating coordinate system, i.e., a magnetization current Im and a torque current It.

The torque current It and the magnetization current Im are sent to a torque-voltage control section 21 and a magnetization-voltage control section 22, respectively. A torque-current command value It* is inputted from a target-torque-current determination section 24 into the torque-voltage control section 21. The torque-voltage control section 21 performs a PI calculation such that a deviation between the torque-current command value It* and a present torque current It becomes 0, thereby determining a torque-voltage command value Vt*. The target-torque-current determination section 24 is a velocity controller, and performs a PI calculation to determine the torque-current command value It* which is such that a deviation between an angular-velocity command value ω*, inputted from an outside of a vector controller 11, and a present angular velocity ac of a motor M becomes zero.

A magnetization-current command value Im* is inputted from a target-magnetization-current determination section 26 into the magnetization-voltage control section 22. The magnetization-voltage control section 22 performs a PI calculation such that a deviation between the magnetization-current command value Im* and the present magnetization current Im becomes 0, thereby determining a magnetization-voltage command value Vm*. A target-magnetization-current determination section 26 determines, by a PI calculation, a magnetization-current command value Im* which is such that a deviation between a target-output-voltage value Vout*, which is sent from a target-output-voltage determination section 27, and a calculated value Vout of the present output voltage becomes zero.

The present output voltage Vout of the inverter 10 is determined by an output voltage calculator 30 from the torque-voltage command value Vt* and the magnetization-voltage command value Vm*. The torque-voltage command value Vt* and the magnetization-voltage command value Vm* are sent to a velocity calculator 31, where the present angular velocity ω of a rotor is determined. This angular velocity ω is inputted into the target-torque-current determination section 24, the target-output-voltage determination section 27, and an integrator 33. The integrator 33 integrates the angular velocity ω to determine the phase θ of the rotor. The phase θ is inputted into the stationary-to-rotational coordinate transformation section 18 and a rotational-to-stationary coordinate transformation section 35.

The magnetization-voltage command value Vm* and the torque-voltage command value Vt* are inputted into the rotational-to-stationary coordinate transformation section 35, where the magnetization-voltage command value Vm* and the torque-voltage command value Vt* on a rotating coordinate system are transformed, based on the phase θ, into a torque-voltage command value and a magnetization-voltage command value on a stationary coordinate system. Further, the torque-voltage command value and the magnetization-voltage command value on the stationary coordinate system are transformed by a two-to-three phase transformation section 36 into voltage command values Vu*, Vv*, Vw* of three phases (i.e., u-phase, v-phase, w-phase). As described above, the inverter 10 generates a voltage in accordance with the voltage command values Vu*, Vv*, Vw*.

The sensorless vector control illustrated in FIG. 19 is a control method which estimates a position of a rotor from a feedback motor current, without using a position sensor.

However, in the above-described sensorless vector control, the magnetization-voltage control section 22, which is a PI controller, calculates the value Vm*, which is used in the velocity calculator 31, which is another PI controller, for calculating the angular velocity co in such a manner that the value Vm* becomes 0. Accordingly, the control by the magnetization-voltage control section 22 interferes with the control by the velocity calculator 31, making it difficult to perform stable control. Specifically, the value Vm*, which is calculated by the magnetization-voltage control section 22 in order to make zero (0) the deviation between the magnetization-current command value Im* and the present magnetization current Im, is inputted as a control object into the velocity calculator 31. Therefore, it is difficult to calculate a stable gain value.

CITATION LIST Patent Literature

Patent document 1: Japanese laid-open patent publication No. 2012-50285

SUMMARY OF INVENTION Technical Problem

The present invention has been made in view of the problem in the prior art. It is therefore an object of the present invention to provide a driving apparatus for an electric motor which can eliminate interference between PI controllers and can achieve stable vector control.

Solution to Problem

In order to achieve the object, the present invention, in one aspect, provides a driving apparatus for an electric motor, comprising: an inverter; a current detector configured to detect an output current of the inverter; and a vector controller configured to transform the output current, detected by the current detector, into a torque current and a magnetization current, and to control the torque current and the magnetization current, wherein the vector controller comprises: a three-to-two phase transformation section configured to transform three-phase currents, detected by the current detector, into two-phase currents; a stationary-to-rotational coordinate transformation section configured to transform the two-phase currents on a stationary coordinate system, which have been transformed by the three-to-two phase transformation section, into a torque current and a magnetization current on a rotating coordinate system; a torque-voltage control section configured to determine a torque-voltage command value based on a deviation between a torque-current command value and the torque current; a magnetization-voltage output section configured to output 0 as a magnetization-voltage command value; a rotational-to-stationary coordinate transformation section configured to transform the torque-voltage command value and the magnetization-voltage command value on a rotating coordinate system into a torque-voltage command value and a magnetization-voltage command value on a stationary coordinate system; a two-to-three phase transformation section configured to transform the torque-voltage command value and the magnetization-voltage command value, which have been transformed by the rotational-to-stationary coordinate transformation section, into three-phase voltage command values; a velocity calculator configured to calculate an angular velocity of a rotor of the electric motor from the magnetization current, a magnetization-current command value, and the torque-voltage command value; a target-torque-current determination section configured to determine the torque-current command value based on a deviation between the angular velocity and an angular-velocity command value; a target-output-voltage determination section configured to determine a target-output-voltage value from the angular velocity of the rotor; and a target-magnetization-current determination section configured to determine the magnetization-current command value based on a deviation between the torque-voltage command value and the target-output-voltage value.

In a preferred embodiment of the present invention, the target-output-voltage determination section stores a V/co pattern in advance, the V/o pattern indicating a relationship between the target-output-voltage value and the angular velocity, and the target-output-voltage determination section is configured to determine the target-output-voltage value from the angular velocity according to the V/o pattern.

In a preferred embodiment of the present invention, the relationship between the target-output-voltage value and the angular velocity, indicated by the V/co pattern, is a relationship in which a ratio between the target-output-voltage value and the angular velocity is constant.

In a preferred embodiment of the present invention, the relationship between the target-output-voltage value and the angular velocity, indicated by the V/o pattern, is a relationship in which a ratio between the target-output-voltage value and the angular velocity is expressed by a square reduction curve.

In a preferred embodiment of the present invention, the target-output-voltage determination section stores a plurality of V/ω patterns in advance, each of the plurality of V/ω patterns indicating a relationship between the target-output-voltage value and the angular velocity, and the target-output-voltage determination section is configured to determine the target-output-voltage value from the angular velocity according to one V/ω pattern selected from the plurality of V/ω patterns.

In a preferred embodiment of the present invention, the relationship between the target-output-voltage value and the angular velocity, indicated by the V/ω pattern, is a relationship in which the target-output-voltage value is kept constant at a rated voltage of the electric motor after the target-output-voltage value has reached the rated voltage.

In a preferred embodiment of the present invention, the relationship between the target-output-voltage value and the angular velocity, indicated by the V/ω pattern, is a relationship in which the target-output-voltage value is kept constant at a rated output voltage of the inverter after the target-output-voltage value has reached the rated output voltage.

In a preferred embodiment of the present invention, the target-magnetization-current determination section stores therein a lower limit value in advance, and is configured to output the lower limit value as the magnetization-current command value when the angular velocity is not more than a predetermined value.

In a preferred embodiment of the present invention, the target-output-voltage determination section stores therein a lower limit value in advance, and is configured to output the lower limit value as the target-output-voltage value when the angular velocity is not more than a predetermined value.

Advantageous Effects of Invention

According to the present invention, stable control can be achieved by setting the magnetization-voltage command value at 0 and fixing the output voltage to a T-axis. Further, one of PI controllers can be eliminated as compared to the conventional sensorless vector control shown in FIG. 19. Therefore, the control operation becomes easier.

BRIEF DESCRIPTION OF DRAWINGS

FIG. 1 is a block diagram showing a driving apparatus according to an embodiment of the present invention;

FIG. 2 is a schematic diagram showing a detail of an inverter shown in FIG. 1;

FIG. 3A is a diagram showing an equivalent circuit of a synchronous motor;

FIG. 3B is a diagram showing an equivalent circuit of a synchronous motor;

FIG. 4 is a diagram showing an output current Iout and an output voltage Vout of the inverter, each of which is expressed as a vector;

FIG. 5 is a diagram showing a control block which determines a target value of a torque current;

FIG. 6A is a diagram showing a relationship between current vector on dq-axes and current vector on MT-axes at a maximum operating efficiency;

FIG. 6B is a diagram showing Vout as a vector corresponding to Iout shown in FIG. 6A;

FIG. 7A is a diagram showing a relationship between current vectors Iout, Iq, It, Im when Id<0;

FIG. 7B is a diagram showing a voltage vector Vout corresponding to the current vector Iout shown in FIG. 7A;

FIG. 8A is a diagram showing a relationship between current vectors Iout, Iq, It, Im when Id>0;

FIG. 8B is a diagram showing a voltage vector Vout corresponding to the current vector Iout shown in FIG. 8A;

FIG. 9 is a diagram showing a control block which determines a magnetization-current command value Im* which is a target value of magnetization current Im;

FIG. 10A is a diagram showing an exemplary Vout*/ω relationship expressed as a linear function;

FIG. 10B is a diagram showing an exemplary Vout*/ω relationship expressed as a square reduction curve;

FIG. 11 is a diagram illustrating an example in which a magnetization-current command value in a low-frequency range is boosted;

FIG. 12 is a diagram illustrating an example in which a load, coupled to a motor, is provided with a torque meter, and illustrating compensation for a decrease in the efficiency of the motor;

FIG. 13 is a graph showing a relationship between torque signal and bias voltage;

FIG. 14 is a diagram illustrating an example in which a pump as a load is coupled to a motor, the pump being further coupled to a pipe which is provided with a flow meter, and illustrating compensation for a decrease in the efficiency of the motor;

FIG. 15 is a graph showing a relationship between flow rate and bias voltage;

FIG. 16 is a diagram illustrating an example of compensating for an efficiency of an entirety of a system including the inverter;

FIG. 17 is a graph showing a relationship between output current of the inverter and bias voltage;

FIG. 18 is a diagram showing a variation of the driving apparatus according to an embodiment of the present invention; and

FIG. 19 is a control block diagram illustrating a conventional sensorless vector control.

DESCRIPTION OF EMBODIMENTS

Embodiments of the present invention will now be described with reference to the drawings.

FIG. 1 is a block diagram showing a driving apparatus according to an embodiment of the present invention. This driving apparatus is an inverter device (or power conversion device) for driving a motor M. As shown in FIG. 1, the driving apparatus is constituted by a plurality of elements including an inverter 10 and a vector controller 11. Specifically, the driving apparatus includes the inverter 10 for generating a voltage to be supplied to the motor M, the vector controller 11 for determining a voltage command value for the inverter 10, and a current detector (or an ammeter) 12 for detecting an electric current supplied from the inverter 10 to the motor M.

FIG. 2 is a schematic diagram showing a detail of the inverter 10 shown in FIG. 1. The inverter 10 is basically constituted by an inverter circuit 10A as a power converter, and a gate driver 10B for driving the inverter circuit 10A. In the inverter circuit 10A, three pairs of upper and lower arms are connected in parallel between a positive line P and a negative line N. DC power (e.g., DC power from a DC power source obtained by full-wave rectification of a commercial power source) is supplied to the positive line P and the negative line N. An antiparallel circuit, composed of switching elements (IGBT) S1 to S6 and diodes D1 to D6, is incorporated in the upper and lower arms of each phase. A symbol C1 represents a capacitor. The inverter circuit 10A is composed of the switching elements S1 to S6, the diodes D1 to D6, and the capacitor C1. The gate driver 10B is configured to drive the switching elements S1 to S6 of the inverter circuit 10A so as to generate a voltage in accordance with the voltage command value sent from the vector controller 11.

The current detector 12 measures three-phase currents Iu, Iv, Iw supplied from the inverter 10 to the motor M. The measured values of the three-phase currents are amplified by a gain adjuster 15, and are then inputted into the vector controller 11. The gain adjuster 15 may be omitted. Measuring of the three-phase currents Iu, Iv, Iw may comprise firstly measuring the currents of any two phases, and then determining the remaining current from an equation: Iu+Iv+Iw=0. The vector controller 11 generates three-phase voltage command values Vu*, Vv*, Vw*, based on the three-phase currents Iu, Iv, Iw and an angular-velocity command value inputted from the outside. Further, the vector controller 11 generates PWM signals corresponding to the three-phase voltage command values Vu*, Vv*, Vw*, and sends the PWM signals to the gate driver 10B. The gate driver 10B generates gate-drive PWM signals based on the PWM signals corresponding to the three-phase voltage command values Vu*, Vv*, Vw*. The six switching elements S1 to S6 are operated (on/off) based on the gate drive-PWM signals. The inverter 10 thus generates a voltage based on the three-phase voltage command values from the vector controller 11, and applied the voltage to the motor M.

A basic operation of the vector controller 11 is as follows. The three-phase output currents of the inverter 10, detected by the current detector 12, are transformed into two-phase currents (vectors) on a rotating coordinate system. When one axis of the rotating coordinate system coincides with a direction of a magnetic flux of a magnet of the motor M, the other axis is perpendicular to the magnetic flux of the magnet of the motor M. Therefore, controlling of the current vector on the axis perpendicular to the magnetic flux of the magnet of the motor M can achieve controlling of the torque of the motor M. Specifically, PI control is performed to determine two-phase voltage command values that can eliminate a deviation between the transformed two-phase currents values and their corresponding target values. The determined two-phase voltage command values on the rotating coordinate system are transformed into three-phase voltage command values on a stationary coordinate system. Then, the PWM signals, corresponding to the voltage command values of each phase, are generated, and the PWM signals are sent to the gate driver 10B of the inverter 10. The vector controller 11 may be comprised of a CPU (central processing unit) or a dedicated processing device.

The vector controller 11 will now be described in detail with reference to FIG. 1. The three-phase currents Iu, Iv, Iw, detected by the current detector 12, are sent to a three-to-two phase transformation section 17, where the three-phase currents Iu, Iv, Iw on a stationary coordinate system are transformed into two-phase currents on the stationary coordinate system. The two-phase currents on the stationary coordinate system are sent to a stationary-to-rotational coordinate transformation section 18, where the two-phase currents are transformed, based on a phase θ, into two-phase currents on a rotating coordinate system, i.e., a magnetization current Im and a torque current It.

The torque current It and the magnetization current Im are sent to a torque-voltage control section 21 and a velocity calculator 31, respectively. A torque-current command value It* is inputted from a target-torque-current determination section 24 into the torque-voltage control section 21. The torque-voltage control section 21 performs a PI calculation so that a deviation between the torque-current command value It* and the present torque current It becomes 0, thereby determining a torque-voltage command value Vt*. The target-torque-current determination section 24 is a velocity controller, and performs a PI calculation to determine the torque-current command value It* which can eliminate a deviation between an angular-velocity command value ω*, inputted from the outside of the vector controller 11, and the present angular velocity ω of the motor M.

A target-magnetization-current determination section 26 is configured to determine, by a PI calculation, a magnetization-current command value Im* which can eliminate a deviation between a target-output-voltage value Vout* and the present output voltage Vout (=Vt*). The target-output-voltage value Vout* is sent from a target-output-voltage determination section 27 (which will be described later in detail).

The magnetization-current command value Im* is inputted from the target-magnetization-current determination section 26 into the velocity calculator 31. A phase synchronizing circuit (or phase-locked loop) may be used as the velocity calculator 31. The velocity calculator 31 performs a PI calculation so as to eliminate a deviation between the magnetization-current command value Im* and the present magnetization current Im, and performs signal processing with the torque-voltage command value Vt* to determine the present angular velocity a of a rotor. This angular velocity en is inputted into the target-torque-current determination section 24, the target-output-voltage determination section 27, and an integrator 33. The integrator 33 integrates the angular velocity ω to determine the phase θ of the rotor. The phase θ is inputted into the stationary-to-rotational coordinate transformation section 18 and a rotational-to-stationary coordinate transformation section 35.

The torque-voltage control section 21 and a magnetization-voltage output section 23 are coupled to the rotational-to-stationary coordinate transformation section 35. The magnetization-voltage output section 23 outputs 0 as a magnetization-voltage command value Vm* to the rotational-to-stationary coordinate transformation section 35. This magnetization-voltage output section 23 is not a PI control unit, and is configured to simply output 0 as the magnetization-voltage command value Vm*. Moreover, the magnetization-voltage output section 23 is not directly connected to the velocity calculator 31, and therefore no interference of control operations occurs between the magnetization-voltage output section 23 and the velocity calculator 31.

The magnetization-voltage command value Vm* [0] and the torque-voltage command value Vt* are inputted into the rotational-to-stationary coordinate transformation section 35, where the magnetization-voltage command value Vm* and the torque-voltage command value Vt* on a rotating coordinate system are transformed, based on the phase θ, into a torque-voltage command value and a magnetization-voltage command value on a stationary coordinate system. Further, the torque-voltage command value and the magnetization-voltage command value on the stationary coordinate system are transformed by a two-to-three phase transformation section 36 into voltage command values Vu*, Vv*, Vw* of three phases (u-phase, v-phase, w-phase). As described above, the inverter 10 generates a voltage in accordance with the voltage command values Vu*, Vv*, Vw*.

A description will now be given of a case in which the vector controller 11 controls a permanent magnet-type synchronous motor. When a d-axis coincides with a direction of a magnetic flux generated by a permanent magnet of a rotor, and a q-axis is perpendicular to the d-axis in a dq rotating coordinate system, an equivalent circuit of the synchronous motor can be given as shown in FIGS. 3A and 3B. In FIGS. 3A and 3B, R represents a winding resistance, Ld represents an inductance in a d-axis direction, Lq represents an inductance in a q-axis direction, ω represents an angular velocity, and E represents an induced voltage.

FIG. 3A shows the equivalent circuit when an electric current Id flows in the d-axis direction, and FIG. 3B shows the equivalent circuit when an electric current Iq flows in the q-axis direction. Referring to FIGS. 3A and 3B, voltage equations are expressed as follows:

Vd=Id·R+pLdId−ωLqIq  (1)

Vq=Iq·R+pLqIq+ωLdId+E  (2)

where p represents a temporal differentiation (d/dt). A symbol j shown in FIGS. 3A and 3B represents an imaginary unit. When the interference components jωLqIq and jωLdId are expressed on the dq-axes (motor axes), the vector direction is changed and the symbol j comes off; therefore, the symbol j does not appear in the equations (1) and (2). In the equations (1) and (2), the induced voltage E is the product of the angular velocity co and an interlinkage magnetic flux Ψ generated by the permanent magnet.

Because of the inductance components (L), a phase lag occurs in the output voltage Vout of the inverter 10 with respect to the output current Iout of the inverter 10. FIG. 4 is a diagram showing the output current Iout and the output voltage Vout of the inverter 10, each expressed as a vector. In FIG. 4, a T-axis is an axis that coincides with a phase of an output voltage Vout-i when the motor is in an ideal control state, and an M-axis is an axis perpendicular to the T-axis. A phase difference β exists between the MT-axes and the dq-axes. In this embodiment, the vector control of the motor is performed using a voltage Vt and a current It on the T-axis and a voltage Vm and a current Im on the M-axis.

The MT-axes are axes for use in controlling of the inverter 10, and are therefore herein called inverter axes. Since Ψ, Ld, Lq, etc. are needed to determine the phase difference β, particular motor constants are necessary. In this regard, this embodiment employs an approach which can control It and Im without using such particular motor constants.

In this embodiment, the T-axis is used as a reference axis, and therefore the voltage component Vm* of the M-axis is made 0. A voltage Vt is applied to the T-axis and a voltage Vm is applied to the M-axis, and the control is performed such that the output current Iout coincides with the q-axis.

FIG. 5 shows a control block which determines a target value of the torque current It. A target value of the torque current, i.e., a torque-current command value It*, is generated by the target-torque-current determination section 24. An angular-velocity command value ω* and the present angular velocity ω are inputted into the target-torque-current determination section 24, which determines the torque-current command value It* for eliminating a deviation between these two values ω* and ω. The angular-velocity command value ω* is a desired angular velocity required for the motor M, and is inputted from the outside of the vector controller 11 into the target-torque-current determination section 24. The present angular velocity ω is given by the velocity calculator 31. The velocity calculator 31 performs a PI calculation so as to eliminate the deviation between the value Im*, determined by the target-magnetization-current determination section 26, and the present magnetization current Im. Further, the velocity calculator 31 determines an estimated angular velocity by processing a signal of the torque-voltage command value Vt*. This estimated angular velocity is used as the present angular velocity ω.

If the angular-velocity command value ω* is larger than the present angular velocity ω (i.e., if ω*>ω), the target-torque-current determination section 24 outputs a larger torque-current command value It* so as to increase the torque and the velocity. In contrast, if the angular-velocity command value ω* is lower than the current angular velocity ω (i.e., if ω*<ω), the target-torque-current determination section 24 outputs a smaller torque-current command value It* so as to decrease the torque and the velocity.

A process of determining the magnetization-current command value Im*, which is a target value of the magnetization current Im, will now be described. For ease of descriptions, in the following embodiment, an SPM (Surface Permanent Magnet) motor is used as the synchronous motor. In the SPM motor, the highest operating efficiency is achieved when the output current Iout from the inverter 10 flows perpendicularly to the d-axis. It is therefore desirable to control the output current of the inverter 10 such that the current Id on the d-axis becomes 0. FIG. 6A shows a relationship between current vector on the dq-axes and current vector on the MT-axes when the highest motor operating efficiency is achieved.

The output voltage Vout of the inverter 10 can be determined from the equations (1) and (2) as follows:

Vout(→)=Vd(→)+Vq(→)  (3)

Vout=Id·R+pLdId−ωLqIq+Iq·R+pLqIq+ωLdId+ωΨ  (4)

where a symbol (→) represents a vector.

When the motor M is in a stable operation, the output current is in the form of a neat sine wave. During the stable operation, the coordinate-transformed currents It and Im change little and can be regarded as being in a steady state. Therefore, the differential term in the equation (4) is negligible. Accordingly, the equation (4) can be expressed as follows:

$\begin{matrix} \begin{matrix} {{Vout} = {{{Id} \cdot R} - {\omega \; {LqIq}} + {{Iq} \cdot R} + {\omega \; {LdId}} + {\omega\Psi}}} \\ {= {{{Id} \cdot R} + {{Iq} \cdot R} + {\omega \left( {{LdId} - {LqIq} + \Psi} \right)}}} \end{matrix} & (5) \end{matrix}$

Further, since the vector Iout is the synthesis of the vector Id and the vector Iq, the equation (5) can be expressed as follows:

Vout=Iout·R+ω(LdId−LqIq+Ψ)  (6)

Since Id is zero (i.e., Id=0) in the state shown in FIG. 6A, Iq is equal to Iout (Iq=Iout). Therefore, the equation (6) can be expressed as follows:

Vout=Iq·R−ωLqIq+ωΨ  (7)

FIG. 6B is a diagram showing Vout as a vector corresponding to Iout shown in FIG. 6A. Since FIG. 6A shows an ideal state when Id is 0, the output voltage at that time is referred to as an ideal output voltage Vout-i. The T-axis coincides with the direction of the vector of the ideal output voltage Vout-i.

FIG. 7A shows a relationship between Iout, Iq, It, and Im in a case where a phase lead of the output current Iout occurs with respect to the current Iq, i.e., when Id<0. Under a condition that the torque current It is controlled at the same magnitude as that of FIG. 6A based on the torque-current command value It*, a tip of the vector Iout lies on a straight line, which is perpendicular to the T-axis and extends through a tip of the vector It. Accordingly, the vector Iq is smaller than that in the ideal state shown in FIG. 6A. The vector of the corresponding voltage Vout is as shown in FIG. 7B. Since Id is smaller than zero, i.e., Id<0, IdR is a leftward vector, and ωLdId is a downward vector. Because of the presence of these vectors and also because of the smaller Iq, the output voltage Vout is smaller than the ideal output voltage Vout-i shown by dotted line (see FIG. 6B). At this time, the current Im on the M-axis is smaller than the current Im in the ideal state shown in FIG. 6A.

FIG. 8A shows a relationship between Iout, Iq, It, and Im in a case where a phase lag of the output current Iout occurs with respect to the current Iq, i.e., when Id>0. Under a condition that the torque current It is controlled at the same magnitude as that of FIG. 6A based on the torque-current command value It*, Iq is larger than that in the ideal state shown in FIG. 6A. The vector of the corresponding voltage Vout is as shown in FIG. 8B. Since Id is larger than zero, i.e., Id>0, IdR is a rightward vector, and ωLdId is an upward vector. Because of the presence of these vectors and also because of the larger Iq, the output voltage Vout is larger than the ideal output voltage Vout-i shown by dotted line (see FIG. 6B). At this time, the current Im on the M-axis is larger than the current Im in the ideal state shown in FIG. 6A.

The followings can be seen from FIGS. 6A through 8B regarding the magnetization current Im. When an actual output voltage Vout is smaller than an ideal output voltage Vout-i, the magnetization current Im is increased to cause the phase lag of the output current Iout, so that the output voltage Vout can approach the ideal output voltage Vout-i. In contrast, when an actual output voltage Vout is larger than an ideal output voltage Vout-i, the magnetization current Im is decreased to cause the phase lead of the output current Iout, so that the output voltage Vout can approach the ideal output voltage Vout-i. In this manner, the magnetization-current command value Im* can be determined by determining a target output voltage for a particular operating state, and determining the deviation between the target output voltage and an actual output voltage.

In the above-described SPM motor, a magnetic flux generated by a winding of a motor stator receives a uniform magnetoresistance of a permanent magnet. Accordingly, the d-axis inductance Ld is equal to the q-axis inductance Lq. In a case of an IPM (Interior Permanent Magnet) motor, a magnetic flux in the d-axis direction receives a magnetoresistance of a permanent magnet, while a magnetic flux in the q-axis direction passes through only an iron core. Therefore, a difference exists between the d-axis inductance Ld and the q-axis inductance Lq. Accordingly, the highest driving efficiency is achieved when the output current Iout has a certain degree of phase lead from the q-axis. However, an angle of this phase lead cannot be calculated without particular motor constants.

However, the relationships shown in FIGS. 7A through 8B hold true also for an IPM motor. Thus, increasing Im will result in an increase in Vout with respect to the ideal output voltage Vout-I, and decreasing Im will result in a decrease in Vout. Therefore, also in an IPM motor, the magnetization-current command value Im* can be determined by determining a target output voltage for a particular operating state, and determining the deviation between the target output voltage and an actual output voltage.

In a case of an induction motor, unlike a synchronous motor, it is necessary to supply a large amount of magnetization current Id in order to generate a magnetic flux, and an inductive power E is generated in the d-axis which is perpendicular to the magnetic flux generated. However, the relationships shown in FIGS. 7A through 8B hold true also for the induction motor. Thus, increasing Im will result in an increase in Vout with respect to the ideal output voltage Vout-I, and decreasing Im will result in a decrease in Vout. Therefore, the magnetization-current command value Im* can be determined by determining a target output voltage for a particular operating state, and determining the deviation between the target output voltage and an actual output voltage.

In this embodiment, a target-output-voltage value Vout*, corresponding to an ideal output voltage Vout-i, is predetermined. A magnetization-current target value Im* is determined based on a deviation between the target-output-voltage value Vout* and the present output voltage. A V/ω pattern, which indicates a relationship between target-output-voltage value Vout* and angular velocity co, is stored in advance in the vector controller 11, as described later in more detail. The vector controller 11 determines the target-output-voltage value Vout*, corresponding to the present angular velocity co, according to the V/co pattern, and further determines the magnetization-current target value based on the deviation between the target-output-voltage value Vout* and the present output voltage Vout.

FIG. 9 shows a control block which determines the magnetization-current command value Im* which is a target value of the magnetization current Im. As shown in FIG. 9, the magnetization-current command value Im* is determined by inputting the target-output-voltage value Vout* and the present output voltage Vout into the target-magnetization-current determination section 26. The present output voltage Vout can be obtained by synthesizing signals of voltage command values Vm*, Vt* on the MT-axes, obtained as a result of the vector control (Vout=√(Vm*²+Vt*²)). In this embodiment, a command voltage is determined using the T-axis as a reference axis. The T-axis is one of the MT-axes which are inverter axes. In this embodiment, 0 is inputted as Vm*. Therefore, the inverter output voltage is located on the T-axis: Vout=Vt*. When Vt*>Vout*, the target-magnetization-current determination section 26 outputs a larger Im* so as to cause the phase lag of the output current Iout, whereas when Vt*<Vout*, the target-magnetization-current determination section 26 outputs a smaller Im* so as to cause the phase lead of the output current Iout.

As shown in FIG. 1, the torque-current command value It* is inputted into the torque-voltage control section 21. As described above, the torque-voltage control section 21 calculates the torque-voltage command value Vt* based on the deviation between the present torque current It and the torque-current command value It*. As described above, the magnetization-voltage command value Vm* is 0. In this manner, the vector control can be performed using T-axis vectors on the MT-axes which are the inverter axes.

The target-output-voltage value Vout* is outputted from the target-output-voltage determination section 27, and is inputted into the target-magnetization-current determination section 26. The target-output-voltage determination section 27 determines the target-output-voltage value Vout* based on the present angular velocity ω. More specifically, the V/ω pattern, which indicates a relationship between target-output-voltage value Vout* and angular velocity ω, is stored in advance in the target-output-voltage determination section 27. The V/ω pattern defines a correlation between angular velocity ω and target-output-voltage value Vout*. This V/ω pattern is used to determine a target-output-voltage value Vout* corresponding to the present angular velocity ω of the rotor. The V/ω pattern is stored as a function or table data which indicates a relationship between target-output-voltage value Vout* and angular velocity ω. Based on the V/ω pattern, the target-output-voltage determination section 27 determines a target-output-voltage value Vout* corresponding to the present angular velocity ω. A frequency F can be determined from an angular velocity ω using the known formula ω=2πF. Therefore, it is also possible to store a V/F pattern, which indicates a relationship between target-output-voltage value Vout* and frequency F, in the target-output-voltage determination section 27.

The relationship between target-output-voltage value Vout* and angular velocity ω may be a relationship in which a ratio between Vout* and m is constant or, in the case of driving a pump or fan in which a load torque is proportional to the square of the rotational speed of a motor, the ratio between Vout* and ω may be expressed by a square reduction curve that follows square reduced torque characteristics. The V/ω pattern can be established from a rated voltage and a rated frequency of the motor M according to the same method as a conventional V/F control.

In order to maximize the motor efficiency, it is desirable to make the target-output-voltage value Vout* coincide with an ideal output voltage Vout-i. However, it is possible to control the motor M so long as the target-output-voltage value Vout* does not significantly deviate from the ideal output voltage Vout-i. Unlike the conventional V/F control, the driving apparatus of this embodiment can avoid a loss of synchronism of the rotor by feeding back the output current of the inverter 10 to the vector controller 11. Furthermore, the feedback of the output voltage Vout to the target-magnetization-current determination section 26 enables the highly-accurate and highly-efficient control operation, compared to the mere V/F control.

In order to establish a linear function in which the ratio Vout*/ω is constant, it is only necessary to know the rated voltage and the rated frequency (or the rated rotational speed) of the motor M as shown in FIG. 10A, while no other particular motor constants are needed. As shown in FIG. 10B, also in the case of expressing the ratio between the target-output-voltage value Vout* and the angular velocity ω by a square reduction curve, a decrement can be determined arbitrarily if the rated voltage and the rated frequency of the motor M are known.

Field-weakening control may be performed in the driving apparatus of this embodiment. Specifically, when the frequency (or the rotational speed) of the motor M exceeds the rated frequency of the motor M, the magnetization current Im is lowered so that the output voltage of the inverter 10 is kept at the rated voltage of the motor M. This operation can increase the rotational speed of the motor M while suppressing the output voltage of the inverter 10. In the V/ca patterns shown in FIGS. 10A and 10B, the target-output-voltage value Vout* is kept constant at the rated voltage of the motor M after the target-output-voltage value Vout* has reached the rated voltage of the motor M. Specifically, in a range over an angular velocity corresponding to the rated frequency of the motor M, the target-output-voltage value Vout* is kept at the rated voltage of the motor M. If an upper limit of the output voltage of the inverter 10, calculated from a DC link voltage, is lower than the rated voltage of the motor M, the target-output-voltage value Vout* is kept at the upper limit of the output voltage of the inverter 10.

The target-output-voltage determination section 27 may store a plurality of V/ω patterns each indicating a relationship between target-output-voltage value Vout* and angular velocity ω. In that case, one V/ω pattern is selected from the plurality of V/ω patterns by a setting operation in a not-shown input section. The target-output-voltage determination section 27 determines a target-output-voltage value Vout* from an angular velocity co according to the selected V/ω pattern. For example, the target-output-voltage determination section 27 may store, as the plurality of V/ω patterns, a V/ω pattern in which the ratio Vout*/ω is constant and a V/ω pattern in which the ratio Vout*/ω is expressed by a square reduction curve, so that one V/ω pattern appropriate for the type of load coupled to the motor M can be selected.

It is possible in this embodiment to boost the torque in a low-frequency range. In general, the output current of the inverter 10 is low in a low-motor frequency (rotational speed) range, and therefore it is difficult to control the motor. In view of this, as shown in FIG. 11, it is preferred to set a lower limit of the magnetization-current command value Im*, shown by dashed-dotted line, in a range in which the angular velocity of the motor M is equal to or lower than a predetermined value, and to boost the magnetization-current command value Im* in this low-frequency range. In the example shown in FIG. 11, when the angular velocity of the rotor of the motor M is not more than ω1, the target-magnetization-current determination section 26 outputs a pre-stored lower limit value as the magnetization-current command value Im* shown by solid line. When the angular velocity is more than ω1, on the other hand, the target-magnetization-current determination section 26 calculates a magnetization-current command value Im* which is shown by dotted line and obtained by the PI control, and outputs the resultant value as the magnetization-current command value Im* shown by solid line. In this manner, the torque boost in the low-motor speed range can be effected by thus compensating for the magnetization-current command value Im* in the low-frequency range. In FIG. 11, the line graph indicating the lower limit value of the magnetization-current command value Im* is inclined. This is because a high command value Im* may lead to over-excitation and low efficiency. In order to avoid such over-excitation and to perform quick control with an appropriate command value, the lower limit value of the magnetization-current command value Im* is decreased in accordance with an increase in the angular velocity, thereby making the command value Im* small.

A lower limit value may be provided on the target-output-voltage value Vout*, instead of the magnetization-current command value Im*. In that case, when the angular velocity is equal to or lower than a predetermined value, the target-output-voltage determination section 27 outputs a pre-stored lower limit value as the target-output-voltage value Vout*. On the other hand, when the angular velocity is higher than the predetermined value, the target-output-voltage determination section 27 outputs the target-output-voltage value Vout* determined from the V/o pattern. Also in this case, as with the example shown in FIG. 11, the lower limit value of the target-output-voltage value Vout* is decreased in accordance with an increase in the angular velocity so that quick control can be performed with an appropriate command value.

The above-described torque boost in the low-frequency range may be performed with selected one of the magnetization-current command value Im* and the target-output-voltage value Vout*. More specifically, the above-discussed lower limit value may be provided on both the magnetization-current command value Im* and the target-output-voltage value Vout*, and either the lower limit value of the magnetization-current command value Im* or the lower limit value of the target-output-voltage value Vout* may selectively be outputted from the target-magnetization-current determination section 26 or the target-output-voltage determination section 27. In the case where the lower limit value of the magnetization-voltage command value Vm* is selected, it is preferred to set an upper limit value on the magnetization-current command value Im* in order to prevent a generation of an overcurrent upon over-excitation due to an excessive magnetization-voltage command value Vm*.

In this embodiment, the target-output-voltage value Vout* is determined from the angular velocity ω in the target-output-voltage determination section 27. This target-output-voltage value Vout*, outputted from the target-output-voltage determination section 27, is not always equal to an ideal output voltage. According to the present invention, it is possible to compensate for a decrease in the motor efficiency due to the difference between the target-output-voltage value Vout* and an ideal output voltage in the following manner.

FIG. 12 is a diagram illustrating an example of compensation for a decrease in the efficiency of the motor M in a case in which a load 41, coupled to a motor M, is provided with a torque meter 42. The vector controller 11 is illustrated without describing its details; only the target-output-voltage determination section 27 and its output are illustrated. An angular-velocity command value ω* and a torque signal outputted from the torque meter 42 are inputted into a bias-voltage determination section 43, and a bias voltage is outputted from the bias-voltage determination section 43. The bias voltage is added to a target-output-voltage value Vout* outputted from the target-output-voltage determination section 27, and the resulting value is inputted into the target-magnetization-current determination section 26 (see FIG. 1). The bias voltage can have a positive value or a negative value.

When there is no change in the angular-velocity command value ω, the bias-voltage determination section 43 increases or decreases the bias voltage so as to maximize the torque detected by the torque meter 42. FIG. 13 is a graph showing a relationship between torque signal and bias voltage. In the example illustrated in FIG. 13, the torque signal reaches its maximum when the bias voltage is −10V. The bias-voltage determination section 43 compares torque signals before and after the increase and the decrease in the bias voltage, and determines whether to increase or decrease the bias voltage. When the angular-velocity command value ω* changes, the bias-voltage determination section 43 returns the bias voltage to 0. In this manner, the bias-voltage determination section 43 increases or decreases the bias voltage so as to maximize the torque until the angular-velocity command value ω* changes.

In general, a calculation cycle for the angular-velocity command value ω* is longer than a cycle of the vector control. For example, the angular-velocity command value ω* is calculated at 100-ms intervals, while the cycle of the vector control (i.e., a cycle of determining the target-output-voltage value Vout*) is 1 ms. In this case, there are at least 100 chances to increase or decrease the bias voltage while the angular-velocity command value ω* is constant. The cycle of the increase or the decrease in the bias voltage may be set to be equal to or longer than the cycle of the vector control. For example, in the above case, the bias voltage may be increased or decreased every 5 ms.

FIG. 14 is a diagram illustrating an example of compensation for a decrease in the efficiency of the motor M in a case in which a pump P as a load is coupled to the motor M and a pipe, coupled to the pump P, is provided with a flow meter 52. FIG. 15 is a graph showing a relationship between flow rate and bias voltage. The example illustrated in FIG. 14 differs from the example illustrated in FIG. 12 in that not the torque signal but a flow rate signal outputted from the flow meter 52 is inputted into the bias-voltage determination section 43, and that the bias voltage is increased or decreased so as to maximize the flow rate. The other constructions and operations of this embodiment shown in FIG. 14 are the same as those of the embodiment shown in FIG. 12.

With use of a sensor (i.e., the torque meter 42, or the flow meter 52) for detecting the state of the load coupled to the motor M, the control can be performed at a further increased motor efficiency by increasing or decreasing the bias voltage, to be added to the target-output-voltage value Vout*, so as to maximize the load state.

It is also possible to perform the control not for compensating for the motor efficiency itself but for increasing the efficiency of the inverter, thereby compensating for the efficiency of the entire system. The embodiments illustrated in FIGS. 12 and 14 are directed to the control for achieving the maximum efficiency point of the motor. However, an operation at the maximum efficiency point of the motor is not always the most efficient operation for the entire system including the inverter, etc. Thus, instead of achieving the maximum torque point of the motor, it is possible to maximize the efficiency of the inverter by increasing or decreasing the bias voltage, to be added to the target-output-voltage value Vout*, so as to minimize the inverter output current.

FIG. 16 is a diagram illustrating an example in which such control is performed. FIG. 17 is a graph showing a relationship between inverter output current and bias voltage. The example illustrated in FIG. 16 differs from the examples illustrated in FIGS. 12 and 14 in that not the signal which indicates the state of the load coupled to the motor M but a signal which indicates the output current of the inverter 10 is inputted into the bias-voltage determination section 43, and that the bias voltage is increased or decreased so as to minimize the output current of the inverter 10. The signal of the output current of the inverter 10, to be inputted into the bias-voltage determination section 43, may be a signal from a sensor 12 which detects the output current of the inverter 10.

Alternatively, the bias voltage may be controlled so as to minimize the inverter output power, instead of the inverter output current. The output power of the inverter 10 can be calculated from the output current and the output voltage of the inverter 10. Therefore, a sensor 40 for detecting the output voltage of the inverter 10 may be provided as shown by two-dot chain lines in FIG. 16, and signals from the sensors 12, 40 that detect the output current and the output voltage may be inputted into the bias-voltage determination section 43. Instead of the signal from the sensor 40, a command voltage value used in the vector controller 11 may be used as the output voltage of the inverter 10.

FIG. 18 is a diagram showing the driving apparatus according to another embodiment of the present invention. In this embodiment, the output voltage is not determined from the voltage command values Vm*, Vt*. Specifically, the three-phase output voltages of the inverter 10 are directly detected by the voltage detector 40. The detected three-phase output voltages are sent to the output voltage calculator 30, where the output voltage Vout of the inverter 10 is determined. As with the above-described embodiment, the output voltage Vout obtained is inputted into the target-magnetization-current determination section 26.

The previous description of embodiments is provided to enable a person skilled in the art to make and use the present invention. Moreover, various modifications to these embodiments will be readily apparent to those skilled in the art, and the generic principles and specific examples defined herein may be applied to other embodiments. Therefore, the present invention is not intended to be limited to the embodiments described herein but is to be accorded the widest scope as defined by limitation of the claims.

INDUSTRIAL APPLICABILITY

The present invention is applicable to a driving apparatus which performs vector control based on an inverter output current.

REFERENCE SIGNS LIST

-   -   10 inverter     -   11 vector controller     -   12 current detector     -   17 three-to-two phase transformation section     -   18 stationary-to-rotational coordinate transformation section     -   21 torque-voltage control section     -   22 magnetization-voltage control section     -   23 magnetization-voltage output section     -   24 target-torque-current determination section     -   26 target-magnetization-current determination section     -   27 target-output-voltage determination section     -   30 output voltage calculator     -   31 velocity calculator     -   33 integrator     -   35 rotational-to-stationary coordinate transformation section     -   36 two-to-three phase transformation section     -   40 voltage detector 

What is claimed is:
 1. A driving apparatus for an electric motor, comprising: an inverter; a current detector configured to detect an output current of the inverter; and a vector controller configured to transform the output current, detected by the current detector, into a torque current and a magnetization current, and to control the torque current and the magnetization current, wherein the vector controller comprises: a three-to-two phase transformation section configured to transform three-phase currents, detected by the current detector, into two-phase currents; a stationary-to-rotational coordinate transformation section configured to transform the two-phase currents on a stationary coordinate system, which have been transformed by the three-to-two phase transformation section, into a torque current and a magnetization current on a rotating coordinate system; a torque-voltage control section configured to determine a torque-voltage command value based on a deviation between a torque-current command value and the torque current; a magnetization-voltage output section configured to output 0 as a magnetization-voltage command value; a rotational-to-stationary coordinate transformation section configured to transform the torque-voltage command value and the magnetization-voltage command value on a rotating coordinate system into a torque-voltage command value and a magnetization-voltage command value on a stationary coordinate system; a two-to-three phase transformation section configured to transform the torque-voltage command value and the magnetization-voltage command value, which have been transformed by the rotational-to-stationary coordinate transformation section, into three-phase voltage command values; a velocity calculator configured to calculate an angular velocity of a rotor of the electric motor from the magnetization current, a magnetization-current command value, and the torque-voltage command value; a target-torque-current determination section configured to determine the torque-current command value based on a deviation between the angular velocity and an angular-velocity command value; a target-output-voltage determination section configured to determine a target-output-voltage value from the angular velocity of the rotor; and a target-magnetization-current determination section configured to determine the magnetization-current command value based on a deviation between the torque-voltage command value and the target-output-voltage value.
 2. The driving apparatus according to claim 1, wherein the target-output-voltage determination section stores a V/ω pattern in advance, the V/ω pattern indicating a relationship between the target-output-voltage value and the angular velocity, and the target-output-voltage determination section is configured to determine the target-output-voltage value from the angular velocity according to the V/ω pattern.
 3. The driving apparatus according to claim 2, wherein the relationship between the target-output-voltage value and the angular velocity, indicated by the V/ω pattern, is a relationship in which a ratio between the target-output-voltage value and the angular velocity is constant.
 4. The driving apparatus according to claim 2, wherein the relationship between the target-output-voltage value and the angular velocity, indicated by the V/ω pattern, is a relationship in which a ratio between the target-output-voltage value and the angular velocity is expressed by a square reduction curve.
 5. The driving apparatus according to claim 2, wherein the target-output-voltage determination section stores a plurality of V/ω patterns in advance, each of the plurality of V/ω patterns indicating a relationship between the target-output-voltage value and the angular velocity, and the target-output-voltage determination section is configured to determine the target-output-voltage value from the angular velocity according to one V/ω pattern selected from the plurality of V/ω patterns.
 6. The driving apparatus according to claim 2, wherein the relationship between the target-output-voltage value and the angular velocity, indicated by the V/ω pattern, is a relationship in which the target-output-voltage value is kept constant at a rated voltage of the electric motor after the target-output-voltage value has reached the rated voltage.
 7. The driving apparatus according to claim 2, wherein the relationship between the target-output-voltage value and the angular velocity, indicated by the V/ω pattern, is a relationship in which the target-output-voltage value is kept constant at a rated output voltage of the inverter after the target-output-voltage value has reached the rated output voltage.
 8. The driving apparatus according to claim 1, wherein the target-magnetization-current determination section stores therein a lower limit value in advance, and is configured to output the lower limit value as the magnetization-current command value when the angular velocity is not more than a predetermined value.
 9. The driving apparatus according to claim 1, wherein the target-output-voltage determination section stores therein a lower limit value in advance, and is configured to output the lower limit value as the target-output-voltage value when the angular velocity is not more than a predetermined value. 